Tunable Orbital Angular Momentum System

ABSTRACT

This system and method of for providing a tunable orbital angular momentum system for providing higher order Bessel beams comprising: an acousto-optical deflector configured to receive an input beam, deflect a first portion of the input beam a first deflection angle relative to an axis of propagation and along an optical axis and deflect a second portion of the input beam a second deflection angle relative to the optical axis; a line generator disposed along the optical angle for receiving the first portion and the second portion of the input beam and provide an elliptical Gaussian mean; a log-polar optics assembly disposed along the optical angle for receiving the elliptical Gaussian beam and wrapping the elliptical Gaussian beam with an asymmetric ring; and, a Fourier lens configured to receive the wrapped elliptical Gaussian beam.

RELATED APPLICATIONS

This application is a continuation of U.S. patent application Ser. No.16/725,293 filed Dec. 23, 2019 which claims priority on U.S. ProvisionalPatent Application 62/784,202 titled filed Dec. 21, 2018, all of whichare incorporated by reference.

STATEMENTS REGARDING FEDERALLY SPONSORED RESEARCH

This invention was made with government support under Federal contractsN00014-16-1-3090 and N00014-17-1-2779 awarded by the Office of NavalResearch. The government has certain rights in the invention.

BACKGROUND OF THE INVENTION 1) Field of the Invention

This system is a novel technique for generating higher order Besselbeams integrated in time.

2) Description of the Related Art

In modern computing, communications, data processing and informationtechnologies, the calculations speed, processing times, storage capacityand speed for data retrieval continue to rapidly improve. However, suchimprovements are limited by physical restrictions such as how fastinformation can move from one place to another. Transmissions speeds arelimited by the number bits of information that can be transmitted usinga single photon in a light beam having an orbital angular momentum (OAM)that is not zero. Generally, the number of orthogonal states of theorbital angular momentum of a photon determines the number of bits thatcan be carried by the photon.

One technique for OAM mode switching uses spatial light modulators(SLM). However, this technique and device has a very limited switchingspeed resulting in disadvantages over the present system. While digitalmicro-mirror devices (DMD) can boost switching speeds up to tens of kHz,which is comparable with the switching speed of a direct OAM modeemitter, the DMD micro-mirror pitch limits the spatial resolution and isonly acceptable for lower optical power applications. Further, the modeemitter is limited to only tuning integer OAM modes. Fractional OAMmodes, also referred to as non-integer, continuous, successive, andrational modes are advantageous but not presently provided with DMDtechnologies.

It would also be beneficial if there were fractional OAM Bessel beamsthat could form any number of orthogonal subsets of OAM modes whichcould be advantageous for optical communications, including in-flightoptical security applications. Further, fractional OAM Bessel beams canpreserve the non-diffracting properties that integer OAM beams possess.This property is advantageous for beam propagation applications,including propagation through turbulence and turbid environments. Inaddition, fractional OAM modes generated by a synthesis ofLaguerre-Gaussian (LG) modes can have advantageous structural stabilityon propagation to the far field. Previously, a long coherence lengthlaser source was needed to ensure different OAM modes would interfereproperly. However, disadvantages are present with long coherence lengthlaser sources so that there is a need for the optical path lengthdifference to be small between simultaneously generated beams withdifferent OAM.

The growing interest in properties, including angular and polarizedproperties, of optical beams as new applications are being consideredfor this technology. The ability to quickly switch between OAM modes isadvantageous to this effort and for new applications of this technology.

It is an object of the present system to provide for improvements intechnologies including communication from classical to quantumapplications, optical manipulation of particles, beam shaping, laserbeam machining, microscopy, microlithography, direct energy,filamentation, as well as sensing through turbulence in air andunderwater environments.

It is another object of the system to provide for the tunablecapabilities of present system to improve optical transmissions invarious conditions, including environments that change slowly such asturbulence.

It is an object of the present system to provide for a superposition ofdriving frequencies that result in multiple OAM modes being generatedsimultaneously.

It is an object of the present invention to provide for a system toimprove communications (e.g. high bandwidths, high data rates, minimalabsorption, bandwidth scalability, etc.) and seeks to increase thebandwidth of a communication system along with giving added security andencryption with the OAM charge numbers.

It is an object of the present invention to provide for a system toimprove imaging as OAM topological charge numbers can propagate betterin turbulent environments (e.g., underwater, turbid environments, etc.),especially when a tunable system can scan through the charge numbers toidentify a desirable mode on a time scale faster than the changes in theenvironmental conditions.

BRIEF SUMMARY OF THE INVENTION

The above objectives are accomplished by providing an optical beam withfast and continuously-tunable orbital angular momentum and havepotential applications in classical and quantum optical communications,sensing, and in the study of beam propagation through turbulence. Thistunable orbital angular momentum system can generate optical beams usingan AOD that can wrap elliptically-shaped Gaussian beams with linearphase tilt to provide a ring. The system can be used with an opticalsource that can be continuous wave and/or pulsed. The optical source canbe encoded with information in terms of a time signal and can becomposed of a single wavelength or multiple wavelengths. The system cantransmit single or multiple coherent beams with different OAMtopological charge numbers.

This system can include the use of an AOD in conjunction with log-polartransformation optics and provides for fast and continuous tuning of theorbital angular momentum (OAM) topological charge number of the outputbeams. The system generates beams with integer and fractionaltopological charge numbers. This system can include an acousto-opticdeflector to add a linear phase ramp to an optical beam that can bewrapped into an azimuthal phase. The AOD in conjunction with thelog-polar optics assembly results in a system that can be used at highpower, with fast and continuous OAM mode tuning.

The system herein can provide for a fast-tunable OAM generation systemand method that can utilizes an optical geometric transformation knownas the log-polar transform. The acousto-optical deflector (AOD) is afast modulation device used for stable phase modulation and beamshaping. Bessel beams generated using an AOD array and a cylindricalaxisymmetric AOD have been provided using this system. In this system, anovel technique for OAM switching and tuning using an AOD in conjunctionwith a log-polar coordinate transformation system is provided. In oneconfiguration, the maximum mode switching speed for the experimentalsetup can be measured on the order of 400 kHz, which is determined bythe acoustic velocity of the crystal as well as the beam diameter. For adifferent AOD and a reduced beam size, this speed can reach tens of MHzwith sub-microsecond response time, a distinctive improvement over theprior art.

In one configuration, an RF signal is applied to the AOD to produce atraveling wave in a crystal. The frequency of the acoustic signalcorresponds to the angle of the 1^(st) order diffraction relative to the0^(th) order. The system is designed around this angle to producespecific OAM topological charge numbers. As the frequency of the appliedsignal is varied, the deflection angle of the 1^(st) order changesaccordingly. Each frequency corresponds to a specific deflection angleand therefore, a unique OAM charge number. Since the frequency can becontrolled with a continuous range, the generated OAM charge numbers canalso be generated in a precise and continuous fashion.

In one configuration, the AOD can support a superposition of acousticsignals, producing multiple output beams with different OAM chargenumbers. The different OAM modes leaving the system will then coherentlyinterfere.

An AOD can be used to continuously tune the deflection angle of anoutput optical beam. Because the AOD has a high damage threshold, andcan therefore be used in high power laser systems for beam deflectingand laser pulse generation, the integration of an AOD with log-polartransformation optics provides for high power and directed energyrelated applications not previously possible in the prior art.

The tunable orbital angular momentum system can include an acousto-opticdeflector adapted to receive an input beam deflected along an opticalaxis when a voltage is applied to the acousto-optic deflector whereinthe acousto-optic deflector outputs a first output beam having a firstdeflection beam and a second deflection beam wherein the firstdeflection beam is in a tilted phase relative to an axis of propagation;a line generator disposed along the optical axis adapted to receive thefirst output beam and provide a second output beam having an ellipticalbeam; and, a log-polar optics assembly disposed along the optical axisadapted to receive the second output beam and adapted to transform thesecond output beam into a third output beam having an asymmetricannular-distribution and to provide a fourth output linear phase wrappedinto an asymmetric ring with azimuthal orbital angular momentum phase.

The input beam can include a flat wavefront. The log-polar opticsassembly can be adapted to provide an elliptical Gaussian beam having anazimuthal orbital angular momentum phase. The second output beam can bean elliptical beam with an elongated length, a suppressed height and aphase tilt along a horizontal direction specific to an applied acousticfrequency. A Fourier lens can be included and adapted to receive thefourth output prior to the fourth output being provided. The log-polaroptics assembly can include a first log-polar optic and a secondlog-polar optic cooperatively associated to map the second output beamto an asymmetric ring profile. The first log-polar optic and the secondlog-polar optic can be cooperatively associated to map the second outputbeam to a phase-corrector adapted to correct a phase distortionintroduced by a wrapper. The input beam can be a Gaussian input.

The system can include a deflection angle defined by the firstdeflection beam and the second deflection beam that is continuouslytunable by adjusting a frequency of an acoustic signal of theacousto-optic deflector. The system can include a first 4-f linegenerator adapted to image the first deflection beam into a line shapebeam's linear phase and a second 4-f line generator adapted to elongatea circular input beam into the input beam. The line generator can beadapted to shape the first deflection beam and the second deflectionbeam of the input beam into an elliptical Gaussian beam using a firstlens and a second lens. The acousto-optical deflector can be is adaptedto add a linear phase gradient to the input beam. The line generator canbe adapted to elongate the first deflection beam and the seconddeflection beam of the input beam into an elliptical Gaussian line.

The fourth output can be an optical beam carrying digital data. Thefourth output can be a wrapped elliptical Gaussian beam adapted forsecure digital communication. The fourth output can be a wrappedelliptical Gaussian beam adapted to manage spatial coherence of beamsfor structured light imaging. The acousto-optic deflector can include acrystal adapted as a Q-switch modulators in a solid state laser.

The log-polar optics assembly can be disposed along the optical axis andadapted to receive the second output beam and adapted to transform thesecond output beam into a third output beam having an asymmetricannular-distribution to provide a fourth output linear phase wrappedinto an asymmetric ring with azimuthal orbital angular momentum phasewherein the fourth output includes multiple modes. The multiple modescan be provided by applying a superposition of multiple RF frequencies.The multiple modes can include factional modes.

This system can alco include a log-polar optics assembly adapted toreceive an input beam having an orbital angular momentum and provide afirst output beam; an acousto-optic deflector adapted to receive thefirst output beam and scan through a frequency range and detect chargenumbers associated with the input beam; and, a fiber coupled detectoradapted for receiving the first output beam and determining the orbitalangular momentum modes. The system can include a first telescope adaptedto receive the input beam prior to the input beam being received by thelog-polar optics assembly and a second telescope adapted to receive anoutput beam from the log-polar optics assembly and project the outputbeam to the acousto-optic deflector.

BRIEF DESCRIPTION OF THE SEVERAL VIEWS OF THE DRAWINGS

The construction designed to carry out the invention will hereinafter bedescribed, together with other features thereof. The invention will bemore readily understood from a reading of the following specificationand by reference to the accompanying drawings forming a part thereof,wherein an example of the invention is shown and wherein:

FIG. 1 is a schematic of aspects of the system;

FIG. 2 is a diagram of aspects of the system;

FIG. 3 is a diagram of aspects of the system;

FIG. 4 is an illustration of aspects and results of the system;

FIG. 5 shows illustrations of aspects and results of the system;

FIG. 6 shows illustrations of aspects and results of the system;

FIG. 7 shows illustrations of aspects and results of the system;

FIG. 8 shows illustrations of aspects and results of the system;

FIG. 9 is a schematic of aspects of the system;

FIG. 10 is an illustration of aspects and results of the system;

FIG. 11A is an illustration of aspects and results of the system;

FIG. 11B is an illustration of aspects and results of the system;

FIG. 12A is an illustration of aspects and results of the system;

FIG. 12B is an illustration of aspects and results of the system;

FIG. 13 is an illustration of aspects and results of the system;

FIGS. 14A and 14B are illustrations of aspects and results of thesystem; and,

FIGS. 15A and 15B are illustrations of aspects and results of thesystem;

DETAILED DESCRIPTION OF THE INVENTION

To improve speeds of information transmission and communications, atthis invention has the capability of switching or hopping between OAMmodes can significantly increase data transmissions rates. Suchtechnical improvements in computer functionality can provide for theincreased efficiency in computer system and information system as awhole. Further, when using the OAM beams provided for by the presentinvention, switching between different OAM modes can provide fordifferent propagation performances through turbulence environmentthereby improving transition rates. The fast switching between OAM modescan provide for the ability to investigate a wide range of OAM modes.Further, sensing applications can benefit from rapidly tunable OAM thatincludes beam steering through a scattering media, particle manipulationusing three dimensional beams, object rotation detection, temperaturesensing, and motion detection. Therefore, transmission of data can beimproved and customized to the environment dynamically.

With reference to the drawings, the invention will now be described inmore detail. Referring to FIG. 1 , an optical configuration 10 used togenerate OAM modes is shown. In this technique, an input beam 12,Gaussian or otherwise, is passed through an acousto-optic deflector(“AOD”) 14. When a voltage signal with the central frequency of the AODis applied, the 1^(st) order deflection of the Gaussian input is at theBragg condition with the Gaussian beam propagating along the opticalaxis. In this orientation, the Gaussian beam can have a flat wavefrontand the designed system will generate an OAM mode of charge equal tozero, 16 a. When the frequency of the acoustic wave deviates from thiscenter frequency, the beam is instead deflected by some additional angle16 b along the horizontal direction. The deviation away from the Braggcondition results in the 1^(st) order deflection with a tilted phaserelative to the axis of propagation. The output of the AOD is thenpassed through a line generator 18, used as a dual-axis manipulator. Theoutput of the line generator can include an elliptical beam with anelongated length and a suppressed height with a phase tilt along thehorizontal direction specific to the applied acoustic frequency. Theline generator can be an f-type in one embodiment. This elliptical beamthen propagates through log-polar optics assembly 20 that wrap theellipse into an asymmetric annular-distribution. The beam can then passthrough a Fourier lens 22. Overall, this results in an ellipticalGaussian beam with linear phase being wrapped into an asymmetric ringwith azimuthal OAM phase.

Referring to FIG. 2 , the input into the AOD can have a Gaussiandistribution with the diameter of the beam defined as 2_(w) ₀ as shownby 32 a. The momentum vector of incident photon can be {right arrow over(k_(i))}, that of the diffracted photon can be {right arrow over(k_(d))}, and that of the photon can be {right arrow over (K)}.According to the principle of momentum conservation, the momentum vectorof the diffracted photon should be equal to the sum of the momentumvectors of the incident photon and of the acoustic phonon {right arrowover (k_(d))}={right arrow over (k_(i))}+{right arrow over (K)}, asshown in FIG. 3 . The notation {right arrow over (k_(d,0))} and {rightarrow over (k_(d.m) )} is used for the diffracted photon's momentumvector when the far-field beam has charge 0 and m, respectively. The OAMmode index m=I+α is a continuous charge number in which I is the integerpart and α is the fractional part, which is defined as a positive realnumber 0≤α<1. The Bragg angle in FIG. 1 can be represented as

$\begin{matrix}{{{\theta_{B} \cong {\sin\theta_{B}}} = {\frac{❘\overset{\rightarrow}{K}❘}{2{❘\overset{\rightarrow}{k_{l}}❘}} = \frac{\lambda_{0}f_{0}}{2V_{a}}}},} & (1)\end{matrix}$

where λ₀ is the electromagnetic wave Doppler shifted wavelengthscorresponding to the OAM charge 0, V_(a) is the acoustic velocity and f₀is the driving frequency of the AOD that results in the Bragg condition,and can also be the frequency corresponding with charge 0 output. The1^(st) order diffractive angle can be 2θ_(B). By deviating the appliedfrequency away from the Bragg condition, Δf_(m)=|f₀−f_(m)|, where f_(m)is the AOD driving frequencies corresponding with charge m output, thereis a change in the deflection angle of the beam for charge m as

$\begin{matrix}{{{\Delta\theta_{m}} = {{❘{\theta_{m} - \theta_{0}}❘} = {{{❘{\frac{\lambda_{m} \cdot f_{m}}{V_{a}} - \frac{\lambda_{0} \cdot f_{0}}{V_{a}}}❘} \approx \frac{\lambda_{m} \cdot {❘{f_{m} - f_{0}}❘}}{V_{a}}} = \frac{{\lambda_{m} \cdot \Delta}f_{m}}{V_{a}}}}},} & (2)\end{matrix}$

where λ_(m) is the electromagnetic wave Doppler shifted wavelengthscorresponding to the OAM charge m. Since these wavelengths are extremelyclose with each other, differing by femtometers for a 532 nm inputsignal, we can assume λ_(m)≈λ₀. The angle deviation after the linegenerator, Δθ′_(m), will be scaled by the magnification of the 1^(st)4-f system according to

$\begin{matrix}{{{\Delta\theta}^{\prime} = {{\Delta\theta}_{m}\frac{F_{1}}{F_{2}}}},} & (3)\end{matrix}$

where F₁ and F₂ are the focal lengths of the lenses L₁ and FL₁,respectively, in FIG. 1 . According to the paraxial approximation, thisangle deviation corresponds to charge m and can be represented by

$\begin{matrix}{{{{\Delta\theta}_{m}^{\prime} \approx {\tan\left( {\Delta\theta}_{m}^{\prime} \right)}} = \frac{\lambda_{m}m}{2\pi a}},} & (4)\end{matrix}$

where α is the log-polar optics design parameter that scales thetransformed line length in the unwrapping procedure. Combining Eq.(2)-(4) results in an expression for charge in as a function of thefrequency change from the Bragg condition given by

$\begin{matrix}{{m = \frac{2\pi{a\left( {\Delta f_{m}} \right)}F_{1}}{V_{a}F_{2}}}.} & (5)\end{matrix}$

As shown in FIG. 1 , the 1^(st) order deflected beam exiting the AOD isa Gaussian distribution, which can be expressed as

$\begin{matrix}{{U_{{AOD}_{1{st}}}\left( {u,v} \right)} = {{{\exp\left\lbrack {- \frac{\left( {u^{2} + v^{2}} \right)}{w_{o}^{2}}} \right\rbrack}{\exp\left\lbrack {i\left( {{2{\pi\left( {f_{c} + f_{m}} \right)}t} - {\overset{\rightarrow}{k_{d.m} \cdot}\overset{\rightarrow}{r}}} \right)} \right\rbrack}} = {{\exp\left\lbrack {- \frac{\left( {u^{2} + v^{2}} \right)}{w_{o}^{2}}} \right\rbrack}{{\exp\left\lbrack {i\left( {{2{\pi\left( {f_{c} + f_{m}} \right)}t} - {k_{z}z} - {k_{u}u}} \right.} \right\rbrack}.}}}} & (6)\end{matrix}$

where u and v are both Cartesian coordinates, f_(c) is the input laser'scentral frequency, k₂=2π cos(Δθ_(m))/λ_(m) and k_(u)=2πsin(Δθ_(m))/λ_(m)≈2πΔθ_(m)/λ_(m) are the wavenumbers along the z and udirection, and finally (f_(c)+f_(m)) and λ_(m) are the electromagneticwave Doppler shifted frequency and wavelength corresponding to the OAMcharge m. After passing through the AOD 14 (FIG. 1 ), the beam is sentto the line generator to be shaped into an elliptical Gaussiandistribution using lenses L₁, L₂ and L₃ with focal lengths F₁, F₂ andF₃, respectively. The elliptical Gaussian beam now has diameters in bothdimensions, defined as 2w_(v)=2w_(o)F₃/F₂ and 2w_(u)=2w₀F₂/F₁. Theelliptical beam can be expressed as

$\begin{matrix}{{{U_{line}\left( {u,v} \right)} = {{\exp\left\lbrack {- \left( {\frac{u^{2}}{w_{u}^{2}} + \frac{v^{2}}{w_{v}^{2}}} \right)} \right\rbrack}{\exp\left\lbrack {i\left( {{2{\pi\left( {f_{c} + f_{m}} \right)}t} - {k_{z}^{\prime}z} - {k_{u}^{\prime}u}} \right)} \right\rbrack}}},} & (7)\end{matrix}$

where the wavenumber along z direction is k′_(z)=2π cos(Δθ_(m)′)/λ_(m)=2π cos(Δθ_(m)F₁/F₂)/λ_(m), and the wavenumber along udirection is k_(u)′=2πΔθ_(m)′/λ_(m)=m/a.

The elliptical Gaussian beam is then incident on the log-polar optics.The system uses a mapping process that uses two log-polar optics: thewrapper that maps the elliptical Gaussian beam to an asymmetric ringprofile, and the phase-corrector that corrects the phase distortionintroduced by the wrapper. Since the elliptical line has a horizontalGaussian distribution, the system wraps it into an asymmetric ring witha ring radius, ρ₀, defined from the origin to peak intensity locationand width, 2w_(ring), as shown in FIG. 3 . Given the log-polar mappingequation of u=a arctan(y/x)=aϕ, the near-field output from the system isgiven by

$\begin{matrix}{{{U_{near}\left( {\rho,\phi} \right)} = {{\exp\left\lbrack {- \left( {\frac{\left( {\rho - \rho_{0}} \right)^{2}}{w_{ring}^{2}} + \frac{\phi^{2}}{\left( {\beta\pi} \right)^{2}}} \right)} \right\rbrack}{\exp\left\lbrack {i\left( {{{- m}\phi} + {2{\pi\left( {f_{c} + f_{m}} \right)}t} - {k_{z}^{\prime}z}} \right)} \right\rbrack}}},} & (8)\end{matrix}$

where ρ and ϕ are both the radial and azimuthal polar coordinates in thenear-field plane, ρ₀=b exp(−v₀/a) is the wrapped ring's radius definedfrom the origin to peak intensity location, w_(ring)=ρ₀ sin h(w_(v)/a)is the wrapped ring's half width v₀, is the input elliptical Gaussianbeam's offset from the center of the wrapper, w_(v)=w₀F₃/F₂ is the halfwidth of the input elliptical Gaussian beam, a is the log-polar opticsdesign parameter which scales the transformed line length in unwrappingprocedure, b is another log-polar optics design parameter which scalesthe transformed ring size in the wrapping procedure, and β=w₀F₂/(πaF₁)is the ratio of input elliptical Gaussian line's length to the designedinput line length 2πa. The Fourier transform of Eq. (8) can then bederived as

$\begin{matrix}{{{U_{far}\left( {r,\theta} \right)} = {A{\exp\left( {- \frac{r^{2}}{w_{G}^{2}}} \right)}{\exp\left\lbrack {i\left( {{2{\pi\left( {f_{c} + f_{m}} \right)}t} - {k_{z}^{\prime}z}} \right)} \right\rbrack}{\sum_{n = {- \infty}}^{\infty}{B_{n}{\exp\left( {in\theta} \right)}{J_{n}\left( {\frac{2{\pi\rho}_{0}}{\lambda_{m}F}r} \right)}}}}},} & (9)\end{matrix}$

where r and θ are the radial and azimuthal polar coordinates in the farfield plane, A=w_(ring) ²βπ^(5/2) ρ₀/(2λ₀F), w_(G)=λ_(m)F/(πw_(ring)), Fis the focal length of the Fourier lens, B_(n)=(−i)^(n-1)2exp[−β²π²(1+α−n)²/4] Im[erfi(i/β+βπ(1+α−n)/2)], erfi(x)=erf(ix)/i is theimaginary error function, and finally Im(z) gives the imaginary part ofcomplex number z. The far-field of the ring-shaped beam in Eq. (9) isthe combination of a group of Bessel-Gaussian (BG) beams carrying OAM.It can be a weighted linear combination of integer OAM phase carryingnth-order Bessel function of the 1^(st) kind modulated by the sameGaussian envelope. The parameter B_(n) is the weighting or selectionfactor, which distributes the power within the central 2 to 3 modes anddecays rapidly as in approaches positive and negative infinity. Whenα=0, then m=l, meaning an integer charge will be select as n=l, andB_(l) is the maximum value. As a increases, the central weighting factorB_(n)'s maximum value will move from n=l to n=l+1. This meansfractional-charged OAM-carrying BG beams are a linear combination ofinteger BG beams. Considering the α=0 case, the B_(n) parameter has theproperty of

B _(m−k)=(−1)^(k) B _(m+k) ,k=0,1,2, . . .  (10)

The far-field complex amplitude described by Eq. (9) can be rewritten as

$\begin{matrix}{{U_{far}\left( {r,\theta} \right)} = {A{\exp\left( {- \frac{r^{2}}{w_{G}^{2}}} \right)}{{\exp\left\lbrack {i\left( {{m\theta} + {2{\pi\left( {f_{m} + f_{c}} \right)}t} - {k_{z}^{\prime}z}} \right)} \right\rbrack} \cdot \left\{ {{B_{m}{J_{m}\left( \frac{2\pi\rho_{0}r}{\lambda_{m}F} \right)}} + {i\sin\theta\frac{m{\lambda}_{m}F}{{\pi\rho}_{0}r}B_{m + 1}{J_{m}\left( \frac{2\pi p_{0}r}{\lambda_{m}F} \right)}} + {\cos\theta{B_{m + 1}\left\lbrack {{J_{m + 1}\left( \frac{2{\pi\rho}_{0}r}{\lambda_{m}F} \right)} - {J_{m - 1}\left( \frac{2\pi p_{0}r}{\lambda_{m}F} \right)}} \right\rbrack}} + {\sum_{k = 1}^{\infty}\left\{ {{B_{m + {2k} + 1}\left\{ {{{\cos\left( {\left( {{2k} + 1} \right)\theta} \right)}\left\lbrack {{J_{m + {2k} + 1}\left( \frac{2{\pi p}_{0}r}{\lambda_{m}F} \right)} - {J_{m - {2k} - 1}\left( \frac{2{\pi\rho}_{0}r}{\lambda_{m}F} \right)}} \right\rbrack} + {i{{\sin\left( {\left( {{2k} + 1} \right)\theta} \right)}\left\lbrack {{J_{m + {2k} + 1}\left( \frac{2{\pi\rho}_{0}r}{\lambda_{m}F} \right)} + {J_{m - {2k} - 1}\left( \frac{2{\pi\rho}_{0}r}{\lambda_{m}F} \right)}} \right\rbrack}}} \right\}} + {B_{m + {2k}}\left\{ {{{\cos\left( {2k\theta} \right)}\left\lbrack {{J_{m + {2k}}\left( \frac{2{\pi\rho}_{0}r}{\lambda_{m}F} \right)} + {J_{m - {2k}}\left( \frac{2{\pi\rho}_{0}r}{\lambda_{m}F} \right)}} \right\rbrack} + {i{{\sin\left( {2k\theta} \right)}\left\lbrack {{J_{m + {2k}}\left( \frac{\mspace{2mu}{2{\pi\rho}_{0}r}}{\lambda_{m}F} \right)} - {J_{m - {2k}}\left( \frac{2{\pi\rho}_{0}r}{\lambda_{m}F} \right)}} \right\rbrack}}} \right\}}} \right\}}} \right\}}}} & (11)\end{matrix}$

This indicates that these beams are comprised of only one integer OAMphase exp(imθ), and the Bessel term of B_(m)J_(m)(2πp₀r/λ_(m)F)dominates, since B_(m) is the maximum of B_(n). The standing wave termssin θ·mλ_(m)FB_(m+1)J_(m)(2πρ₀r/λ_(m) F)/πρ₀r and cosθ·B_(m+1)[J_(m+1)(2πρ₀r/λ_(m)F)−J_(m−1)(2πρ₀r/λ_(m)F)] contribute to theasymmetric intensity of this group of BG beams. In fact, the rest of theB_(n) factors are really small in comparison with the central term andcontribute minimally to the BG beam, but still in the form of standingwaves.

As can be seen in Eq. (11), a change in β only affects the weightingfactor B_(n). Conceptually, when μ is very small, very little power willbe contained at the edges of the active zone on the log polar elements.When this whole area is wrapped, there will be a highly asymmetric ring.As β approaches 1, the distribution about the wrapped ring becomes moreazimuthally Gaussian. In fact, as β increases beyond 1, the distributionabout the wrapped ring becomes more azimuthally uniform and theweighting factors B_(l±1) decrease, but more of the power will beclipped by the log-polar optic aperture. This results in a lower powerefficiency of the system but higher modal symmetry. Eq. (9) not onlydescribes the distribution of integer charge numbers, but alsofractional charge numbers.

Referring to FIG. 4 , analytic intensity and phase profiles usingsimulation parameters λ=532 nm, β=0.66, w_(ring)=329 μm, ρ₀=850 μm,using 5 central terms, and for the focal length of Fourier lens F=400 mmis shown. Amplitude is shown as 34 with phase shown as 36.Traditionally, the log-polar coordinate transform theory assumes thatthe input is a rectangular shaped beam. This input results in a reducedtranslation efficiency due to the fact that a Fourier transform of arectangular function contains high spatial frequency components.Further, a Gaussian shape produces a Gaussian distribution. In thepresent system, however, an elliptical Gaussian beam can be generatedfrom a Gaussian input resulting in a higher power efficiency compared tothat of a rectangular beam input traditionally used.

In order to produce the log-polar optics assembly 20 (FIG. 1 ), thediffractive elements 20 a and 20 b can be fabricated using aphotolithographic method. Referring to FIG. 5 , one configuration can bemade by fabricating a 6 row×6 column device 24 on a single wafer 26. Inone configuration, the optics can be optimized for the wavelength of 532nm, and have a pixel size of 2 μm×2 μm and 2⁴=16 phase levels. Thedesign parameter a can be 1.8/π mm and b can be 2 mm. The microscopeprofiles of a wrapper and phase-corrector are shown as 28 a and 28 b.Scanning-electron microscopy (SEM) images of the fabricated optics areshown as 30 a and 30 b with magnification of 130 times. The diffractionefficiency of a 4-layer lithographic process diffractive phase elementcan be about 98%. A 99.9% transmission anti-reflection (AR) coating canbe applied on each surface of the log-polar optics that can result inthe mean transmission efficiency of both the wrapper and phase correctorcombined of about 91% with 0.5% standard deviation from charge −10 to10.

In one embodiment, the AOD that can couple up to 70% of the opticalenergy into its 1^(st) diffraction order. This deflection angle iscontinuously tunable by adjusting the frequency of the acoustic signal.The system can apply a 4-f system to image the AOD output deflectionangle into the line shape beam's linear phase and another 4-f system toelongate the circular Gaussian beam into an elliptical Gaussian beam.The elliptical Gaussian beam can be incident upon the wrapper and thencan be mapped into an azimuthally asymmetric ring shaped beam duringpropagation to the phase corrector. After phase correction at the secondoptical element, the ring-shaped beam carrying OAM phase will form a BGbeam in the far-field. One configuration is shown in FIG. 6 . The AOD 14is shown receiving incident light which is then transmitted to a linegenerator, such as the 4-f line generator 15 a in this configuration andon to the log-polar optics 20.

In one configuration, the deflected beam can be generated using a Gooch& Housego AODF 4120-3. This AOD is constructed using a tellurium dioxide(TeO₂) crystal, with a Bragg angle of 2.9°, computed by Eq. (1). Theinput 36 having two deflections, passes through the line generator 18and log polar optics 20 to produce an output beam 38.

In this configuration, the acoustic velocity is 0.65 mm/μs, which can betypical for the shear mode of a TeO₂ crystal. An input beam with adiameter of approximately 1.5 mm can be deflected at a rate ofapproximately 434.8 kHz, corresponding to a measured switching speed of2.3 μs. Higher switching speeds can be achievable by using othermaterials such as quartz and fused silica. The acoustic velocity of suchdevices can be an order of magnitude above the shear-mode TeO₂ devices.By decreasing the beam size through a crystal and with a faster acousticvelocity, switching speeds could be further increased into the tens ofmegahertz. The transmission efficiency of each surface of the 3 opticsin the line generator can be 99%, and the total transmission efficiencyof log-polar optics assembly can be 91%. In one configuration, the1^(st) order diffractive efficiency (DE) of the AOD can be 70% so thatthe total system efficiency is about 60%. Using a 30 mW input power, theoutput BG beam is about 18 mW.

In one configuration, the focal lengths L₁ and L₂ are F₁=50 mm andF₂=100 mm respectively, parameter a=1.8/π mm, and the frequency indexcorresponding to Δm=1 interval is Δf₁=0.36 MHz. A series of rings withdifferent OAM phases are output from the log-polar optics assembly. Thefar-field of this group of ring shape OAM phase carrying beams are BGbeams. The generated BG beams are shown in FIG. 6 . Referring to FIG. 7, a comparison of the radius of the dark vortex to the correspondingcharge numbers as well as driving signal frequencies is shown for boththe experimental and simulated beam profiles. This radius was measuredby finding the inner radial location of the half-maximum amplitude. TheDE of the m=−5 beam is 8.8% lower than the DE of the m=5 beam becausethe deviation away from the Bragg condition that has the highest DE. Thesimulated and experiment results of BG beams central dark area's radiusvary with charge number as well as AOD driving signal's frequency.

The deflection angle of the 1^(st) order AOD output is continuouslytunable as well as the OAM phase. A sample of fractional OAM modesspanning from charge −1.2 to +1.2 in steps of 0.6 is shown in FIG. 8 .Referring to FIG. 8 , generated fractional OAM BG beams as shown as (a)charge −1.2, (b) charge −0.6, (c) charge 0, (d) charge 0.6, and (e)charge 1.2.

This system and method provide for cascading an AOD with log-polaroptics assembly providing for transformation of an optical system torapidly and continuously tune the output OAM mode of a BG beam. Thissystem has the capability of generating tunable fractional OAM modes.The OAM mode can be controlled through the AOD driving frequency, whichcan control the amount of linear tilt to be wrapped into a ring throughthe log-polar transformation.

In one configuration, charge number scans can be defined by an arbitrarywaveform across the acousto-optic deflector. The acousto-optic deflectorcan also be high efficiency and can be configured to withstand highpowers with modulation rates 20× over LC spatial light modulators.

The scalar form of the far-field system described herein has results ina group of asymmetric fractional BG beams. This system provides for afast and continuous OAM carrying BG beam tuning solution.

Referring to FIG. 9 , one configuration is shown for spatialmultiplexing using the system described herein. The charge number can berelated to the fiber input port on the input plane. Further, OAMs can becreated from any two input port locations. The charge number can befixed by fiber spacing on the input array and focal length of the lendsin the present design.

Referring to FIG. 10 , results for the present system with a 1550 nmspectrum with simulated results shown as (a) channel 1, m=2.0; (b)channel 2, m=0.7; (c) channel 3, m=−0.7; and (d) channel 4, m=−2.0 andthe corresponding results shown as (e) to (h). The system herein alsoprovides for a linear phase tilt (which can be the same as shifting thepoint source above and below the optic axis). A phase tilt can beintroduced at the input plane to the system.

Referring to FIG. 11A, shows a single charge number continuous scanning+5 to −5. A coherent combination of conjugate pairs continuous scanning+/−5 to 0 is shown in FIG. 11B.

The benefits of the current system can include that OAM can be used forunderwater communications and the implementation of coherentmultiplexing between OAM states has many applications in maritimesensing. The coherent coupling of OAM modes provides for a modulationscheme that can exploit higher order Poincare sphere for 3D and possibly4D Codes. The beams provided by the system described herein can berealized with a combination of optics, amplitude and phase control forcommunications, sensing and directed energy. Quantum communication andsensing can be improved by using the beams and beam control provided bythis system.

Numeric representations of the system described herein is providedbelow. The near-field output from the system represented by Eq. (8) canbe rewritten as separable functions with respect to only ρ or ϕ terms,

$\begin{matrix}{{U_{near}\left( {\rho,\theta} \right)} = {{P(\rho)}{{\Phi(\phi)}.}}} & (12)\end{matrix}$ $\begin{matrix}{{{P(\rho)} = {\exp\left( {- \frac{\left( {\rho - p_{0}} \right)^{2}}{w_{ring}}} \right)}},} & (13)\end{matrix}$ $\begin{matrix}{{\Phi(\phi)} = {{\exp\left\lbrack {- \frac{\phi^{2}}{\left( {\beta\pi} \right)^{2}}} \right\rbrack}{{\exp\left( {{im}\phi} \right)}.}}} & (14)\end{matrix}$

Since the far field light distribution is the Fourier transform of thenear-field, then

$\begin{matrix}{{U_{far}\left( {r,\theta} \right)} = {{\frac{1}{i\lambda_{0}F}\mathcal{F}\left\{ {U_{near}\left( {\rho,\phi} \right)} \right\}} = {\frac{1}{i\lambda_{0}F}\mathcal{F}{\left\{ {\exp\left( {- \frac{\rho^{2}}{w_{ring}^{2}}} \right)} \right\} \cdot \mathcal{F}}{\left\{ {{\delta\left( {\rho - \rho_{0}} \right)}{\exp\left\lbrack {- \frac{\phi^{2}}{\left( {\beta\pi} \right)^{2}}} \right\rbrack}{\exp\left( {im\phi} \right)}} \right\}.}}}} & (15)\end{matrix}$

As shown in Eq. (15), there are two Fourier transforms that can besolved. Starting with the definition of the polar coordinate Fouriertransform,

$\begin{matrix}{{{U_{far}\left( {r,\theta} \right)} = {\frac{1}{i\lambda_{0}F}{\int_{- \pi}^{\pi}{\int_{0}^{\infty}{{U_{near}\left( {\rho,\phi} \right)}{\exp\left( {{- i}\frac{2\pi}{\lambda_{m}F}\rho r{\cos\left( {\theta - \phi} \right)}} \right)}\rho d\rho d\phi}}}}},} & (16)\end{matrix}$

the term

of in Eq. (15) can be written as,

$\begin{matrix}{{\mathcal{F}\left\{ {{\delta\left( {\rho - \rho_{0}} \right)}\exp\left\{ {- \frac{\phi^{2}}{\left( {\beta\pi} \right)^{2}}} \right\}{\exp\left( {im\phi} \right)}} \right\}} = {\int_{- \pi}^{\pi}{\int_{0}^{\infty}{{\delta\left( {\rho - \rho_{0}} \right)}{\exp\left\lbrack {- \frac{\ \phi^{2}}{({\beta\pi})^{2}}} \right\rbrack}{\exp\left( {im\phi} \right)}{{\exp\left( {{- i}\frac{2\pi}{\lambda_{m}F}\rho r{\cos\left( {\theta - \phi} \right)}\rho d\rho d\phi} \right)}.\ }}}}} & (17)\end{matrix}$

Eq. 17 can be expanded into

$\begin{matrix}{{\exp\left( {{- i}\frac{2\pi}{\lambda_{m}F}\rho r{\cos\left( {\theta - \phi} \right)}} \right)} = {\sum_{n = {- \infty}}^{+ \infty}{\left( {- 1} \right)^{n}{J_{n}\left( {\frac{2\pi}{\lambda_{m}F}\rho r} \right)}{{\exp\left\lbrack {i{n\left( {\theta - \phi} \right)}} \right\rbrack}.}}}} & (18)\end{matrix}$

which allows for Eq. 17 to be rewritten as

$\begin{matrix}{{\mathcal{F}\left\{ {{\delta\left( {\rho - \rho_{0}} \right)}\exp\left\{ {- \frac{\phi^{2}}{\left( {\beta\pi} \right)^{2}}} \right\}{\exp\left( {im\phi} \right)}} \right\}} = {\sum_{n = {- \infty}}^{+ \infty}{\left( {- i} \right)^{n}{\exp\left( {in\theta} \right)}{\int_{0}^{\infty}{{\delta\left( {\rho - \rho_{0}} \right)}{J_{l}\left( {\frac{2\pi}{\lambda_{m}F}\rho r} \right)}\rho d\rho{\int_{- \pi}^{\pi}{{\exp\left\lbrack {{- \frac{\phi^{2}}{\left( {\beta\pi} \right)^{2}}} + {i{\phi\left( {m - n} \right)}}} \right\rbrack}d{\phi.}}}}}}}} & (19)\end{matrix}$

The azimuthal integral can be solved by

$\begin{matrix}{{\int_{- \pi}^{\pi}{{\exp\left\lbrack {{- \frac{\phi^{2}}{({\beta\pi})^{2}}} + {i{\phi\left( {m - n} \right)}}} \right\rbrack}d\phi}} = {{\frac{{- i}{\beta\pi}\sqrt{\pi}}{2}{{\exp\left( {- \frac{({\beta\pi})^{2}\left( {m - n} \right)^{2}}{4}} \right)}\left\lbrack {{{erfi}\left( {\frac{i}{\beta} + \frac{{\beta\pi}\left( {m - n} \right)}{2}} \right)} - {{erfi}\left( {{- \frac{i}{\beta}} + \frac{{\beta\pi}\left( {m - n} \right)}{2}} \right)}} \right\rbrack}} = {{\beta\pi}\sqrt{\pi}{\exp\left( {- \frac{({\beta\pi})^{2}\left( {m - n} \right)^{2}}{4}} \right)}{{{Im}\left\lbrack {{erfi}\left( {\frac{i}{\beta} + \frac{{\beta\pi}\left( {m - n} \right)}{2}} \right)} \right\rbrack}.}}}} & (20)\end{matrix}$

The far field light distribution in Eq. (15) reduces to the finalanalytic terms as given by Eq. (9), in which the Bn term is theweighting term and shifts power between different Bessel terms.Considering the α=0 case, given n=m+k=l+k, k=0, 1, 2 . . .

$\begin{matrix}{B_{n = {l + k}} = {{\left( {- i} \right)^{l + k - 1}2{\exp\left( {- \frac{({\beta\pi})^{2}\left( {l - \left( {l + k} \right)} \right)^{2}}{4}} \right)}{{Im}\left\lbrack {{erfi}\left( {\frac{i}{\beta} + \frac{\beta{\pi\left( {l - \left( {l + k} \right)} \right)}}{2}} \right)} \right\rbrack}} = {\left( {- i} \right)^{l + k - 1}2{{\exp\left( {- \frac{\left( {k\beta\pi} \right)^{2}}{4}} \right)} \cdot {{{Im}\left( {{erfi}\left( {\frac{i}{\beta} - \frac{k\beta\pi}{2}} \right)} \right)}.}}}}} & (21)\end{matrix}$

When using the case where n=m−k=l−k,

$\begin{matrix}{B_{n = {l - k}} = {{\left( {- i} \right)^{l - k - 1}2{\exp\left( {- \frac{l - {\left( {l - k} \right)^{2}\left( {\beta\pi} \right)^{2}}}{4}} \right)}{{Im}\left\lbrack {{erfi}\left( {\frac{i}{\beta} + \frac{\left( {l - {\left( {l - k} \right){\beta\pi}}} \right.}{2}} \right)} \right\rbrack}} = {\left( {- i} \right)^{l - k - 1}2{{\exp\left( {- \frac{\left( {k{\beta\pi}} \right)^{2}}{4}} \right)} \cdot {{{Im}\left( {{erfi}\left( {\frac{i}{\beta} + \frac{k{\beta\pi}}{2}} \right)} \right)}.}}}}} & (22)\end{matrix}$

Since the imaginary error function is an odd function, we have

$\begin{matrix}{B_{n = {l - k}} = {{\left( {- i} \right)^{l - k - 1}2{{\exp\left( {- \frac{\left( {k{\beta\pi}} \right)^{2}}{4}} \right)} \cdot {{Im}\left\lbrack {{erfi}\left( {\frac{i}{\beta} + \frac{k\beta\pi}{2}} \right)} \right\rbrack}}} = {{\frac{\left( {- i} \right)^{l + k - 1}}{\left( {- i} \right)^{2k}}2{{\exp\left( {- \frac{\left( {k{\beta\pi}} \right)^{2}}{4}} \right)} \cdot {{Im}\left( {- {{erfi}\left( {{- \frac{i}{\beta}} - \frac{k{\beta\pi}}{2}} \right)}} \right)}}} = {{\left( {- 1} \right)^{k}\left( {- i} \right)^{l + k - 1}2{{\exp\left( {- \frac{\left( {k{\beta\pi}} \right)^{2}}{4}} \right)} \cdot {{Im}\left( {- {{erfi}\left( {{- \frac{i}{\beta}} - \frac{k{\beta\pi}}{2}} \right)}} \right)}}} = {{\left( {- 1} \right)^{k}\left( {- i} \right)^{l + k - 1}2{{\exp\left( {- \frac{\left( {k{\beta\pi}} \right)^{2}}{4}} \right)} \cdot {{Im}\left( {- {{erfi}\left( \overset{\_}{\frac{i}{\beta} - \frac{k{\beta\pi}}{2}} \right)}} \right)}}} = {{\left( {- 1} \right)^{k}\left( {- i} \right)^{l + k - 1}2{{\exp\left( {- \frac{\left( {k{\beta\pi}} \right)^{2}}{4}} \right)} \cdot {{Im}\left( \overset{\_}{- {{erfi}\left( {\frac{i}{\beta} - \frac{k{\beta\pi}}{2}} \right)}} \right)}}} = {\left( {- 1} \right)^{k}{B_{n = {l + k}}.}}}}}}}} & (23)\end{matrix}$

This system can be a receiver as well as a transmitter. This system canalso be used in reverse so that the system provides for a sensor todetect beams with OAM. Instead of generating specific OAM modescorresponding to the RF driving frequency, the AOD can scan through thefrequency range to detect the OAM charge number of incoming beams. Inthe embodiment, the input beam can enter a first telescope and bedirected into the log polar optics. The beam can enter into a secondtelescope and be directed into the AOD. A fiber detector can thenreceive the beam.

Individual beams with OAM modes of m=0 (left), m=−2 (middle) and m=+2(right) were examined using the system. The results shown in FIG. 13 canindicate a single scan in time of frequencies applied to the AOD thatcorrespond to a scan of OAM modes of m=−4 to m=+4. Because of the speedof the AOD, the change in the OAM mode can be monitored in time as shownin the bottom row of figures, resulting in a dynamic OAM mode sorter.

The acousto-optic deflector can include crystals that can be used asQ-switch modulators in solid state lasers. Since these are usedintracavity, they have a large optical power handling capacity and havetypical damage thresholds on the order of MW/cm². The switching speed ofthe present system can be determined by the acoustic wave velocity inthe AOD and the input beam size. The switching speed of the currentsystem has been demonstrated to be on the order of 400 kHz, which ismuch faster than traditional DMD/SLM systems.

Referring to FIGS. 12A and 12B, the AOD can be driven with a singlefrequency or multiple frequencies. Multiple frequencies that generatecharges +m and −m can be applied to the AOD simultaneously to createcoherently combined OAM modes. The deflection of both charge +m and −mcan be 1^(st) order deflections with slightly different deflectionangles. Information can be encoded onto both the amplitude and relativephase of the coherently coupled OAM modes and mapped to athree-dimensional constellation space. The 3D quadrature amplitudemodulation (QAM) constellation can be based on a higher-order Poincaresphere equivalent for OAM states. In one example of the system, a 532 nmlaser can be used with two coherent OAM charges of m=±2 are generatedafter passing through the system by applying frequencies f+2≈124.28 MHzand f−2≈125.72 MHz simultaneously to the AOD. Two different modulationschemes can be applied to the acoustic cell to control the output beam.A 16-PSK signal and a 512-QAM signal with the modulation rate of 200 kHzare shown in FIGS. 12A and 12B. This system can have advantages directedto improving the spectral efficiency of a communications link. Thissystem can improve upon and advantage to encoding schemes andmultiplexing techniques in both free-space and optical fiber-basedcommunication links. Optical beams can be used as a data carrier forboth free-space and underwater communications.

The system can be adapted to operate at about a 450 nm wavelength sothat the diode amplitude can be controlled by an external signal. TheAOD can be used to produce multiple interfering OAM beamssimultaneously. Due to the traveling wave in the AOD, different OAMbeams can have a small shift in the optical frequency, producing acontinuously changing interference pattern due to the continuous changein phase of the sinusoidal waves on the AOD. The diode amplitude can bepulsed as a method of sampling the output beam similar to a strobelight. If the pulse width is on the order of the rate of change of theinterference pattern, and repeats periodically, in synchronization withthe signal applied to the AOD, the beam profile can be sampled andtemporally controlled.

In one example of the system in operation, the laser source is aThorLabs LP450-SF15 single-mode fiber-pigtailed diode placed in aThorLabs LDM9LP pigtailed driver mount. The output is then polarizedvertically and resized to approximately 3 mm in diameter where it ispassed through the AOD. The output of the AOD is then shaped into a lineapproximately 3 mm by 0.3 mm using a soft aperture. The line is thenpassed through the log-polar optical transformation system after which a400 mm lens is used to image the far field beam profile onto a SpiriconSP300 CCD camera with an integration time of 10 ms and a frame rate of30 Hz. The voltage signals applied to the AOD isV=sin(2πf₁t)+sin(2πf₂t+θ) to generate two different structures as shownin FIGS. 14A and 14B. The first signal has frequencies f1=95.4 MHz andf2=84.6 MHz to create a beam with m=±1 and the second signal hasf1=100.9 MHz and f2=79.1 MHz to create a beam with m=±2 for a beatfrequency of 10.9 MHz and 21.8 MHz respectfully. This rotation farexceeds the framerate of the CCD array and therefore the average imageis collected and appears as a ring. FIGS. 14A and 14B illustrate thetime-averaged signal of the system output for a two-beam combination ofm=±1 and m=±2.

In one example, a 20 ns Gaussian pulse was applied to the diode at arepetition rate of 3 MHz which can be greater than the switching speedof the AOD; limited by the velocity of the acoustic wave and the beamdiameter. The voltage signal applied to the AOD can have the samerepetition rate. The CCD array can integrate with approximately 30,000pulses per frame, timed so that the pulse is synced with the signalapplied to the AOD. This pulse can be coupled with a DC bias currentusing a bias-tee located inside a laser diode mount. The DC bias appliedto the laser diode can be set to about 30 mA and/or a level just abovethe threshold. In conjunction with the pulse and the losses in theoptical system, the output pulse incident on the CCD array can have apeak power of 17 mW. In addition, the relative phase between the twosignals θ can be adjusted to rotate the interference fringes. Theseprofiles are shown in FIGS. 15 a and 15 b . for four different phaselevels. Due to the continuous rotation, the pulse and the AOD signalmust be properly aligned to sample the proper beam combination. FIGS.15A and 15B illustrate a time-averaged signal of the system output witha 20 ns Gaussian amplitude pulse for a two-beam combination of FIG. 15Am=±1 and FIG. 15B m=±2. These images show the expected interferencepattern, where the number of fringes is equal to the difference incharge number. In addition, the apparent rotation angle is proportionalto this difference as can be seen. The FWHM of the pulse isapproximately 12% of the rotation rate for the first case andapproximately 26% for the second. This difference is due to the requiredfrequencies listed above, causing a faster rotation rate for the largerbeams. This indicates that there will still be some blurring of the beamover the pulse which could impact sensing systems. It is understood thatthe above descriptions and illustrations are intended to be illustrativeand not restrictive. It is to be understood that changes and variationsmay be made without departing from the spirit or scope of the followingclaims. Other embodiments as well as many applications besides theexamples provided will be apparent to those of skill in the art uponreading the above description. The scope of the invention should,therefore, be determined not with reference to the above description,but should instead be determined with reference to the appended claims,along with the full scope of equivalents to which such claims areentitled. The disclosures of all articles and references, includingpatent applications and publications, are incorporated by reference forall purposes. The omission in the following claims of any aspect ofsubject matter that is disclosed herein is not a disclaimer of suchsubject matter, nor should it be regarded that the inventor did notconsider such subject matter to be part of the disclosed inventivesubject matter.

What is claimed is:
 1. A tunable orbital angular momentum systemcomprising: an acousto-optic deflector adapted to receive an input beamdeflected along an optical axis when a voltage is applied to theacousto-optic deflector wherein the acousto-optic deflector outputs afirst output beam having a first deflection beam and a second deflectionbeam wherein the first deflection beam is in a tilted phase relative toan axis of propagation; a line generator disposed along the optical axisadapted to receive the first output beam and provide a second outputbeam having an elliptical beam; and, a log-polar optics assemblydisposed along the optical axis adapted to receive the second outputbeam and adapted to transform the second output beam into a third outputbeam having an asymmetric annular-distribution and to provide a fourthoutput linear phase wrapped into an asymmetric ring with azimuthalorbital angular momentum phase wherein the log-polar optics assemblyincludes a first log-polar optic and a second log-polar opticcooperatively associated to map the second output beam to an asymmetricring profile.
 2. The system of claim 1 wherein the input beam includes aflat wavefront.
 3. The system of claim 1 wherein the log-polar opticsassembly is adapted to provide an elliptical Gaussian beam having anazimuthal orbital angular momentum phase.
 4. The system of claim 1wherein the second output beam is an elliptical beam with an elongatedlength, a suppressed height and a phase tilt along a horizontaldirection specific to an applied acoustic frequency.
 5. The system ofclaim 1 including a Fourier lens adapted to receive the fourth outputprior to the fourth output being provided.
 6. The system of claim 1wherein the first log-polar optic and the second log-polar opticcooperatively associated to map the second output beam to aphase-corrector adapted to correct a phase distortion introduced by awrapper.
 7. The system of claim 1 wherein the input beam is a Gaussianinput.
 8. The system of claim 1 including a first telescope adapted toreceive the input beam prior to the input beam being received by thelog-polar optics assembly.
 9. The system of claim 1 including a secondtelescope adapted to receive an output beam from the log-polar opticsassembly and project the output beam to the acousto-optic deflector. 10.A tunable orbital angular momentum system comprising: an acousto-opticdeflector adapted to receive an input beam deflected along an opticalaxis when a voltage is applied to the acousto-optic deflector whereinthe acousto-optic deflector outputs a first output beam having a firstdeflection beam and a second deflection beam wherein the firstdeflection beam is in a tilted phase relative to an axis of propagation;a line generator disposed along the optical axis adapted to receive thefirst output beam and provide a second output beam having an ellipticalbeam; a log-polar optics assembly disposed along the optical axisadapted to receive the second output beam and adapted to transform thesecond output beam into a third output beam having an asymmetricannular-distribution and to provide a fourth output linear phase wrappedinto an asymmetric ring with azimuthal orbital angular momentum phase;and, a deflection angle defined by the first deflection beam and thesecond deflection beam that is continuously tunable by adjusting afrequency of an acoustic signal of the acousto-optic deflector.
 11. Thesystem of claim 10 including a first 4-f line generator adapted to imagethe first deflection beam into a line shape beam's linear phase.
 12. Thesystem of claim 10 including a second 4-f line generator adapted toelongate a circular input beam into the input beam.
 13. The system ofclaim 10 wherein the line generator is configured to shape the firstdeflection beam and the second deflection beam of the input beam into anelliptical Gaussian beam using a first lens and a second lens.
 14. Thesystem of claim 10 wherein the acousto-optical deflector is adapted toadd a linear phase gradient to the input beam.
 15. The system of claim10 wherein the line generator is adapted to elongate the firstdeflection beam and the second deflection beam of the input beam into anelliptical Gaussian line.
 16. A tunable orbital angular momentum systemcomprising: an acousto-optic deflector adapted to receive an input beamdeflected along an optical axis wherein the acousto-optic deflectoroutputs a first output beam having a first deflection beam and a seconddeflection beam; a line generator disposed along the optical axisadapted to receive the first output beam and provide a second outputbeam having an elliptical beam; a log-polar optics assembly disposedalong the optical axis adapted to receive the second output beam andadapted to transform the second output beam into a third output beamhaving an asymmetric annular-distribution to provide a fourth outputlinear phase wrapped into an asymmetric ring with azimuthal orbitalangular momentum phase, wherein the fourth output is a wrappedelliptical Gaussian beam adapted for secure digital communication; and,a Fourier lens adapted to receive the fourth output prior to the fourthoutput being provided.
 17. The system of claim 16 wherein the fourthoutput is an optical beam carrying digital data.
 18. A tunable orbitalangular momentum system comprising: an acousto-optic deflector adaptedto receive an input beam deflected along an optical axis wherein theacousto-optic deflector outputs a first output beam having a firstdeflection beam and a second deflection beam; a line generator disposedalong the optical axis adapted to receive the first output beam andprovide a second output beam having an elliptical beam; a log-polaroptics assembly disposed along the optical axis adapted to receive thesecond output beam and adapted to transform the second output beam intoa third output beam having an asymmetric annular-distribution to providea fourth output linear phase wrapped into an asymmetric ring withazimuthal orbital angular momentum phase; and, wherein the fourth outputis a wrapped elliptical Gaussian beam adapted to manage spatialcoherence of beams for structured light imaging.
 19. The system of claim18 wherein the acousto-optic deflector can include a crystal adapted asa Q-switch modulators in a solid state laser.
 20. A tunable orbitalangular momentum system comprising: an acousto-optic deflector adaptedto receive an input beam deflected along an optical axis wherein theacousto-optic deflector outputs a first output beam having a firstdeflection beam and a second deflection beam; a line generator disposedalong the optical axis adapted to receive the first output beam andprovide a second output beam having an elliptical beam; and, a log-polaroptics assembly disposed along the optical axis adapted to receive thesecond output beam and adapted to transform the second output beam intoa third output beam having an asymmetric annular-distribution to providea fourth output linear phase wrapped into an asymmetric ring withazimuthal orbital angular momentum phase wherein the fourth outputincludes multiple modes; and, wherein the multiple modes are provided byapplying a superposition of multiple RF frequencies.
 21. The system ofclaim 20 wherein the multiple modes include factional modes.
 22. Atunable orbital angular momentum system comprising: a log-polar opticsassembly adapted to receive an input beam having an orbital angularmomentum and provide a first output beam; an acousto-optic deflectoradapted to receive the first output beam and scan through a frequencyrange and detect charge numbers associated with the input beam; and, afiber coupled detector adapted for receiving the first output beam anddetermining the orbital angular momentum modes.